Method for controlling a polyphase converter with distributed energy stores at low output frequencies

ABSTRACT

The invention relates to a method for controlling a multi-phase power converter having at least two phase modules ( 100 ) comprising valve branches (T 1 , . . . , T 6 ) having bipolar subsystems ( 10, 11 ) connected in series, at low output frequencies (f). According to the invention, a target value (u 1  (t), . . . , u 6  (t)) of a valve branch voltage overlaps a common-mode voltage (uCM(t)) such that a sum of two valve branch voltages (u 1  (t), U 2  (t) or U 3  (t), U 4  (t) or U 5  (t), U 6  (t)) of each phase module ( 100 ) equals an intermediate circuit voltage (Ud) of said multi-phase power converter. In this manner a known converter having a triphase power converter comprising distributed energy accumulators on the grid and load side, or merely on the load side, may be utilized as a drive converter, which may start up from the idle state.

The invention relates to a method for controlling a converter with at least two phase modules having an upper and a lower valve branch having in each case two two-pole subsystems connected in series at low output frequencies.

Such a converter with distributed energy stores is known from the publication “Modulares Stromrichterkonzept für Netzkupplungsanwendung bei hohen Spannungen”, by Rainer Marquardt, Anton Lesnicar and Jüml urgen Hildinger” [Modular Converter Concept for System Coupling Application at High Voltages], printed in the conference proceedings of the ETG Conference 2002. In this publication, such a converter is used for a system-side and load-side converter, with these two converters being coupled to one another with distributed energy stores on the DC-voltage side.

FIG. 1 shows in more detail such a converter with distributed energy stores. In accordance with this circuit arrangement, this known converter circuit has three phase modules, which are each denoted by 100. These phase modules 100 are connected electrically conductively on the DC-voltage side in each case to a connection P or N with a positive or negative DC voltage busbar P₀ or N₀. A DC voltage U_(d) is present between these two DC voltage busbars P₀ and N₀. Each phase module 100 has an upper and a lower valve branch T1 or T3 or T5 and 12 or T4 or T6. Each of these valve branches T1 to T6 has a number of two-pole subsystems 10 which are connected electrically in series. In this equivalent circuit diagram, four subsystems 10 are illustrated per valve branch T1, . . . , T6. Each node between two valve branches T1 and T2 or T3 and T4 or T5 and T6 of a phase module 100 forms a connection L1 or L2 or L3 of this phase module 100 on the AC-voltage side.

FIG. 2 shows in more detail an embodiment of a known two-pole subsystem 10. The circuit arrangement shown in FIG. 3 represents a functional equivalent variant. These two subsystems 10 and 11 are described in more detail in DE 101 03 031 A1, which laid-open specification also describes the way in which said subsystems operate.

A further embodiment of a two-pole subsystem 20 is shown in more detail in FIG. 3. This embodiment of the two-pole subsystem 20 is known from DE 10 2005 041 087 A1. The design of this two-pole subsystem 20 and the way in which it operates are described in detail in this laid-open specification, and therefore no explanation in relation to this is necessary at this juncture.

The number of independent energy stores 9 and 29, 30 which are connected in series between a positive connection P and a connection L1 or L2 or L3 of a phase module 100 on the AC-voltage side is referred to as the series operating cycle n. It is advantageous here, but not absolutely necessary, to implement the same series operating cycle n between a connection L1 or L2 or L3 on the AC-voltage side and a negative connection N of a phase module 100. As shown in FIG. 1, each valve branch T1, . . . , T6 of the polyphase converter has four two-pole subsystems 10, which are connected electrically in series. Since these subsystems 10 each have only one independent energy store 9, a series operating cycle of n=4 results. If, instead of these subsystems 10, four subsystems 20 are used as shown in FIG. 2, this results in a series operating cycle n=8 since each subsystem 20 has two independent energy stores 29 and 30.

For the following explanation it is assumed that all of the energy stores 9 of the subsystems 10 of each valve branch T1, . . . , T6 of this polyphase converter are each charged to the same voltage U_(c). A method for charging this energy store 9 is described, for example, in the conference proceedings for the ETG Conference 2002.

The voltages u₁(t), . . . , u₆(t) at the valve branches T1, . . . , T6, also referred to as valve branch voltage u₁(t), . . . , u(t), comprise a DC variable ½U_(d) and an AC voltage variable u₁₀(t), u₂₀(t), u₃₀(t). This AC voltage variable u₁₀(t) or u₂₀(t) or u₃₀(t) has, firstly a frequency and an amplitude of a desired output voltage of the converter. These AC variables u₁₀(t), u₂₀(t) and u₃₀(t) are related to a fictitious mid-point 0 between the two DC voltage busbars P₀ and N₀, as shown in FIG. 1. This results in sinusoidal converter output voltages u₁₀(t), u₂₀(t) and u₃₀(t), wherein the following must apply for the amplitudes of the voltages u₁₀(t), u₂₀(t) and u₃₀(t) related to the mid-point 0: each amplitude of an AC voltage variable u₁₀(t), u₂₀(t) and u₃₀(t) should always be less than half the DC voltage U_(d). The voltage u₁(t) or u₂(t) or u₃(t) or u₄(t) or u₅(t) or u₆(t) of a valve branch T1 or T2 or T3 or T4 or T5 or T6 must therefore always be positive since all of the two-pole subsystems 10 of a valve branch T1, . . . , T6 which are connected in series can generate only a short circuit or a positive voltage at the output terminals X1 and X2 of each two-pole subsystem 10, irrespective of the valve branch current direction in all switching states. Owing to the structure of these two-pole subsystems 10, 11 and 20, negative voltages are not possible. Therefore, the valve voltage u₁(t) or u₂(t) or u₃(t) or u₄(t) or u₅(t) or u₆(t) of each valve branch T1 or T2 or 13 or T4 or 15 or 16 can vary between zero and n times a capacitor voltage U_(c) of the n independent energy stores 9 and, respectively, 29, 30.

FIG. 5 shows a characteristic of the valve branch voltage u₁(t) and of the valve branch current i₁(t) of the valve branch T1 of the phase module 100 of the polyphase converter shown in FIG. 1 in a graph over time t. If the two characteristics are multiplied by one another, the time characteristic of an instantaneous power P_(T1)(t) of this valve branch T1 is produced, which is illustrated in a graph over time t in FIG. 6. If this instantaneous power P_(T1)(t) of the valve branch T1 is integrated over a period of the valve branch voltage u₁(t) (corresponds to the areas below the curved sections of the curve of the instantaneous power P_(T1)(t)), in the steady state the value zero is always reached. This means that the energy stores 9 of the two-pole subsystems 10 in this valve branch T1 in total do not receive or emit any energy. The same also applies to all of the other valve branches T2, . . . ,T6 of the polyphase converter shown in FIG. 1.

It follows from this that the energy content of each energy store 9 of each valve branch T1, . . . , T6 of the polyphase converter shown in FIG. 1 and therefore of this polyphase converter is constant in the steady state. For this reason, these two-pole subsystems 10 and 11 and 20 also do not require an active power feed to the respective DC voltage connections of the energy stores 9 and 29, 30, respectively.

An energy content of each energy store 9 or 29, 30 of the two-pole subsystems 10, 11 and 20, respectively, of each valve branch T1, . . . , T6 is advantageously dimensioned in accordance with the maximum required energy deviation. It is necessary here to take into account the fact that the voltage ripple ΔU which is superimposed on the steady-state voltage mean value in the energy stores 9 and 29,30 should not overshoot a maximum predetermined limit value. This maximum voltage is determined by the dielectric strength of the semiconductor switches and energy stores 9 and 29, 30 which can be switched off and are used in the two-pole subsystems 10, 11 and 20, respectively, and also by means of regulation technology. A decisive factor in the dimensioning of the energy stores 9 and 29, 30 is the output frequency of the polyphase converter shown in FIG. 1. The lower this output frequency is, the greater the energy deviation is per period in the energy store 9 or 29, 30. This means that, for a predetermined voltage ripple ΔU, the required variable of the energy stores 9 and 29, 30 of the two-pole subsystems 10, 11 and 20, respectively, would tend towards infinity in hyperbolic fashion as the frequency decreases up to the DC voltage operating mode (frequency equal to zero).

This relationship between the voltage ripple ΔU and the output frequency f of the polyphase converter shown in FIG. 1 is illustrated in a graph shown in FIG. 7. This graph shows a hyperbolic curve A for the voltage ripple of an energy store (continuous line) and a hyperbolic curve B for the voltage ripple when using three partial energy stores in parallel per energy store 9 or 29, 30, i.e. three times the intermediate-circuit capacitance (dashed line). The hyperbolic curve A shows that, starting from an output frequency f=50 Hz, the voltage ripple ΔU increases substantially as the frequency decreases. If at half the output frequency the voltage ripple ΔU should be equal to the voltage ripple ΔU at the output frequency f=50 Hz, the value of an energy store 9 or 29, 30 of a two-pole subsystem 10, 11 or 20 must be a multiple greater.

The graph in FIG. 8 shows a characteristic of the valve branch voltage u₁(t) with an output frequency f=50 Hz and a characteristic of this valve branch voltage u₁(t) at an output frequency of f=5 Hz over time t. The amplitude of the valve branch voltage u₁(t) at an output frequency f=5 Hz has been decreased corresponding to a u/f characteristic. If a recalculation is performed taking into consideration the corresponding valve branch current in the valve branch T1 of the polyphase converter shown in FIG. 1, an associated instantaneous power P_(T1)(t) at an output frequency f=50 Hz and f=5 Hz is produced. These two characteristics of the instantaneous power P_(T1)(t) of the valve branch T1 are shown in the graph in FIG. 9 over time t. The energy deviation at the output frequency f=5 Hz has risen substantially in comparison with the energy deviation at the output frequency f=50 Hz. In this example illustrated, the energy deviation at f=5 Hz is 25 times greater than at f=50 Hz.

In order to produce the same voltage ripple ΔU as at the output frequency f=50 Hz in this operating point as well (f=5 Hz), the energy store 9 or 29, of the two-pole subsystems 10, 11 or 20 would need to be dimensioned to be a factor of 25 greater.

In order to arrive at a solution which is attractive in terms of size and costs, it is advantageous if the design of the energy stores 9 and 29, 30 of the two-pole subsystems 10, 11 and 20, respectively, of the valve branches T1, . . . , T6 of the polyphase converter shown in FIG. 1 is performed for a rated working point. This means that, in this rated working point, the energy deviation already results in a predetermined maximum permissible voltage ripple ΔU. For operation at low frequencies, i.e. below a rated frequency f_(N), up to purely DC operation (f=0 Hz), as arises when running up drives, the control methods in accordance with the prior art cannot be used for a realistic and competitive design of the energy stores 9 and 29, 30 of two-pole subsystems 10, 11 and 20 used.

The invention is now based on the object of specifying a method for controlling a polyphase converter with distributed energy stores, which enables operation at low output frequencies up to the DC operating mode.

This object is achieved according to the invention by the features of claim 1.

In accordance with the invention, a common mode voltage is superimposed on a setpoint value of all of the valve branch voltages of the polyphase converter with distributed energy stores. Since this superimposed AC voltage simultaneously alters the potentials of all three connections, on the AC-voltage side, of the polyphase converter with distributed energy stores in comparison with the potentials of the DC voltage busbars thereof, this modulated AC voltage is referred to as the common mode voltage. The superimposed common mode voltage ensures that the line-to-line output voltages of the polyphase converter with distributed energy stores remain unaffected.

In an advantageous embodiment of the method according to the invention, the common mode voltage is predefined in such a way that the voltage ripple of all of the energy stores 9 and 29, 30 does not overshoot a predetermined maximum value. As a result, the maximum voltage at the energy stores likewise remains below a predetermined maximum value, which is selected in accordance with the dielectric strength of the semiconductors and energy stores.

In a further advantageous embodiment of the method according to the invention, the common mode voltage is predefined in such a way that in each case a predetermined maximum value for the valve branch currents is not overshot. As a result, on-state losses and switching losses which occur in the semiconductor switches which can be switched off of the two-pole subsystems used are restricted to a value.

In a further advantageous embodiment of the method according to the invention, the amplitude of the common mode voltage is inversely proportional to the rise in the output frequency. This means that this common mode voltage is only effective in a frequency band below a rated frequency.

Further advantageous configurations of the method according to the invention are given in dependent claims 5 to 9.

In order to further explain the invention, reference is made to the drawing, which is used to explain the method according to the invention in greater detail.

FIG. 1 shows a circuit diagram of a known three-phase converter with distributed energy stores,

FIGS. 2 to 4 each show an equivalent circuit diagram of a two-pole subsystem of the converter shown in FIG. 1,

FIG. 5 illustrates a graph over time t of a valve branch voltage and an associated valve branch current, whereas

FIG. 6 illustrates a graph over time t of an instantaneous power corresponding to the valve branch voltage and valve branch current shown in FIG. 5 over time t,

FIG. 7 shows a graph of the voltage ripple as a function of the output frequency of the converter shown in FIG. 1,

FIG. 8 shows a graph over time t of a valve branch voltage of the converter shown in FIG. 1 at an output frequency of 50 Hz and 5 Hz,

FIG. 9 shows a graph over time t of associated instantaneous powers,

FIG. 10 shows a graph over time t of a valve branch voltage at an output frequency f=5 Hz with a common mode voltage which is unequal or equal to zero,

FIG. 11 shows a graph over time t of three valve branch voltages of the converter shown in FIG. 1, in each case with a common mode voltage which is not equal to zero, and

FIG. 12 shows an advantageous embodiment of the three-phase converter shown in FIG. 1.

As has already been described at the outset, the following equations apply to the time characteristics of the valve branch voltages u₁(t), . . . , u₆(t):

u₁(t)˜½·U_(d)−u₁₀(t),

u₂(t)˜½·U_(d)+u₁₀(t),

u₃(t)˜½·U_(d)−u₂₀(t),

u₄(t)˜½·U_(d)+u₂₀(t),

u₅(t)˜½·U_(d)−u₃₀(t),

u₆(t)˜½·U_(d)+u₃₀(t).

This means that each valve branch T1, . . . , T6 at each time always produces half the DC voltage U_(d) between the DC voltage busbars P₀ and N₀ which are common to all of the phase modules 100. A sinusoidal component with a predetermined frequency and a desired amplitude of a converter output voltage u₁₀(t), u₂₀(t) or u₃₀(t), which is related to a fictitious mid-point between the voltage busbars P₀ and N₀, is generally superimposed on this direct current variable.

According to the invention, in each case a common mode voltage u_(CM)(t) is superimposed on these valve branch voltages u₁(t), . . . , u₆(t) in such a way that the line-to-line output voltages continue to be excluded thereby. The following equations then apply to the time characteristics of these valve branch voltages u₁(t), . . . , u₆(t).

u₁(t)˜½·U_(d)−u₁₀(t)+u_(CM)(t),

u₂(t)˜½·U_(d)+u₁₀(t)−u_(CM)(t),

u₃(t)˜½·U_(d)−u₂₀(t)+u_(CM)(t),

u₄(t)˜½·U_(d)+u₂₀(t)−u_(CM)(t),

u₅(t)˜½·U_(d)−u₃₀(t)+u_(CM)(t),

u₆(t)˜½·U_(d)+u₃₀(t)−u_(CM)(t).

The graph in FIG. 10 illustrates a valve branch voltage u₁(t) at an output frequency f=5 Hz with a common mode voltage u_(CM)(t) which is once not equal to zero and is once equal to zero over time t. It can be seen from the signal characteristic of the valve branch voltage u₁(t) with a superimposed common mode voltage u_(CM)(t) which is not equal to zero that this common mode voltage u_(CM)(t) is sinusoidal and the amplitude thereof is dimensioned such that the peak value û₁(t) of the valve branch voltage u₁(t) adheres to an upper boundary condition such that the following applies:

0<u ₁(t)<U _(d)

Since output converter currents i_(L1)(t), i_(L2)(t) and i_(L3)(t), also referred to as load currents i_(L1)(t), i_(L2)(t) and i_(L3)(t), and therefore also the valve branch powers P_(T1)(t), . . . , P_(T6)(t) of each valve branch T1, . . . , T6 during operation at a low output frequency f up to an output frequency f=0 (DC operating mode) in the time characteristic now only have very few zero points, or no zero points at all (FIG. 9), the balancing of the energy stores 9 within a voltage branch T1, . . . , T6 and therefore within an electrical period of a converter output voltage u₁₀(t), u₂₀(t) or u₃₀(t) is now no longer sufficient, in contrast to operation at the rated frequency f_(N) given the same energy store size. The periods in which a respectively constant valve current direction is applied to the valve branches T1, . . . , T6 are too long during operation without any modulated common mode voltage u_(CM)(t). As a result, the energy stores 9 and 29, 30 of the two-pole subsystems 10, 11 and 20 used are discharged or charged excessively, which would result in an impermissibly high voltage ripple ΔU in the two-pole subsystems 10, 11 and 20.

The modulation of a common mode voltage u_(CM)(t) forces the onset of an energy interchange between the subsystems 10, 11 and 20, which are in switching state II (U_(x)=U_(c)), of the phase modules 100 of the polyphase converter shown in FIG. 1 which are connected to the DC voltage busbars P₀ and N₀. If the potentials of the converter output voltages u₁₀(t), u₂₀(t) and u₃₀(t) are in the vicinity of the DC voltage busbar P₀ (FIG. 11), the energy stores 9 and 29, 30 of the subsystems 10, 11 and 20 of the lower valve branches T2, T4, T6 adjust their energy content to one another. If the potential of the converter output voltages u₁₀(t), u₂₀(t) and u₃₀(t) is close to the DC voltage busbar N₀ of the polyphase converter shown in FIG. 1, the energy stores 9 and 29, 30 of the subsystems 10, 11 and 20, respectively of the upper valve branches T1, T3 and T5 adjust their energy content to one another.

This adjustment of the energy contents results in an additional valve branch current, which is part of an existing compensating current. In this case, the energy compensation takes place passively, i.e. without any influence by a superimposed open-loop/closed-loop control system. Furthermore, it is also possible to influence the energy compensation in a targeted manner by active influencing of the valve branch currents. In this case, use is made of the method known from the patent specification 10 2005 045 090.

However, the common mode voltage u_(CM)(t) can be used irrespective of the type of energy compensation (passive or active). It is only possible to limit the energy deviation of the energy stores by compensating currents in such a way that the level of these compensating currents does not result in unfavorable overdimensioning of the semiconductors by virtue of a simultaneous shift, as a result of a common mode voltage u_(CM)(t), in the potentials of the converter output voltages u₁₀(t), u₂₀(t) and u₃₀(t).

The additional valve branch current results in increased on-state losses and switching losses in the semiconductor switches which can be disconnected of the two-pole subsystems 10, 11 and 20 used. As a result, however, more favorable dimensioning of the energy stores of the subsystems 10, 11 and 20 used is achieved, i.e., this disadvantage is considered to be insignificant in comparison with the advantage (more favorable energy store dimensions).

When selecting amplitude, curve form (sinusoidal, trapezoidal, triangular, . . . ) and frequency of the common mode voltage u_(CM)(t), in principle there are considerable degrees of freedom for the design. The following points play an important role in the dimensioning of the common mode voltage u_(CM)(t):

-   -   Advantageously, the maximum rate of change

$\left. \frac{{u_{CM}(t)}}{t} \right|_{\max}$

-   -   of the superimposed common mode voltage u_(CM)(t) is selected         such that it is not necessary for a plurality of energy stores 9         and 29, 30 of the subsystems 10, 11 and 20 used of a valve         branch T1, . . . , T6 to be switched simultaneously in order to         follow the predetermined setpoint value characteristic. As a         result, the advantage of the lower motor insulation capacity as         a result of low sudden voltage change levels in comparison with         converters with a low number of stages would sometimes be given         up again. In addition, low sudden voltage change levels have a         positive effect on the level of the bearing and shaft currents         and therefore increase the life of the drive.     -   The longer the potentials in the vicinity of the connections of         the DC voltage busbar P₀ or N₀ of the polyphase converter shown         in FIG. 1 are kept, the better the energy contents of the energy         stores 9 and 29, 30 of the submodules 10, 11 and 20,         respectively, which are in the switching state II can be matched         to one another. For this reason, a trapezoidal curve         characteristic of the common mode voltage u_(CM)(t) with a         pronounced plateau phase appears to be particularly         advantageous, but not absolutely necessary.     -   The common mode voltage u_(CM)(t) is to be dimensioned such that         the resultant valve branch currents do not overshoot maximum         values to be predefined.     -   The common mode voltage u_(CM)(t) needs to be dimensioned such         that the resultant voltage ripple ΔU in the energy stores 9 and         29, 30 of the subsystems 10, 11 and 20, respectively, used does         not overshoot maximum values to be predefined.

When using the modulation of a common mode voltage u_(CM)(t) according to the invention, it is necessary to ensure when using standard system motors that the maximum line-to-ground voltage u_(LE) at the motor is not overshot in order not to damage the motor insulation. In the case of an ungrounded converter with DC isolation from the feed system by a feed-side transformer, it is generally the case that the potential of the neutral point of the machine winding is in the vicinity of the ground potential owing to the capacitive ratios. By virtue of the clocking of the converter, the potential ratios are shifted automatically in the converter. As a result, once the positive DC voltage busbar P₀ is in the vicinity of the ground potential, and once the negative DC voltage busbar N₀ is in the vicinity of the ground potential. In this case, it may arise at high common mode voltages u_(CM)(t) that the total intermediate circuit voltage U_(d) is present at the machine terminals as line-to-ground voltage U_(LE). In the normal case, the following maximum condition therefore applies for the maximum value û_(LE) is of the line-to-ground voltage u_(LE):

${\hat{u}}_{LE} = {U_{d} = {\frac{2\sqrt{2}}{\sqrt{3}}U_{M}}}$

where U_(M): rms value of the line-to-line motor voltage.

Even higher intermediate circuit voltages U_(d) and therefore higher values for û_(LE) are possible, but result in unfavorable design of the converter.

In the case of standard system motors which are designed for operation directly on the sinusoidal supply system, the maximum permissible value û_(LE) of the line-to-ground voltage U_(LE) is lower by a factor of 2, however:

${\hat{u}}_{LEsystem} = {\frac{\sqrt{2}}{\sqrt{3}}U_{M}}$

In order to solve this problem, it is advantageous to connect the fictitious mid-point of the intermediate circuit to the ground potential. This can take place with the aid of a resistor 40, by means of a capacitor 50 or by means of a parallel circuit comprising a resistor 40 and a capacitor 50, as shown in FIG. 12. As a result, the maximum voltage loading is halved and the maximum line-to-ground voltage at the machine terminals can thus be reduced to the maximum value û_(LEsystem) in the case of a sinusoidal system feed.

By means of this method according to the invention, the converter known from the conference proceedings relating to the ETG Conference 2002, which converter has a three-phase converter with distributed energy stores as shown in FIG. 1 on the system and load side, can be used as a drive converter which can be run up from standstill. In this application it is possible, even at low frequencies up to the DC operating mode of this converter, for the energy stores 9 and 29, 30 of the subsystems 10, 11 and 20 used to be dimensioned in optimum fashion. 

1.-9. (canceled)
 10. A method for controlling a polyphase converter at a low output frequency, the converter comprising at least two phase modules, each phase module having an upper and a lower valve branch, with each of the upper and a lower valve branches each comprising at least two two-pole subsystems connected in series, the method comprising superimposing a common-mode voltage on a setpoint value of a voltage of the upper and lower valve branches such that a sum of the voltages of the upper and lower valve branch of each phase module is equal to an intermediate circuit voltage of the polyphase converter.
 11. The method of claim 10, wherein the common mode voltage is selected so that a resulting voltage ripple does not exceed a predetermined maximum value.
 12. The method of claim 10, wherein the common mode voltage is selected so that resulting valve branch current does not exceed a predetermined maximum value.
 13. The method of claim 10, wherein an amplitude of the common mode voltage is inversely proportional to an increase in the output frequency of the polyphase converter.
 14. The method of claim 10, wherein the common mode voltage is trapezoidal.
 15. The method of claim 10, wherein the common mode voltage is sinusoidal.
 16. The method of claim 10, wherein the common mode voltage is triangular.
 17. The method of claim 10, wherein the common mode voltage is selected such that, for a maximum value for a line-to-ground voltage across terminals of a connected motor, the following condition is met: ${\hat{u}}_{LE} \leq U_{d} \leq {\frac{2\sqrt{2}}{\sqrt{3}}U_{M}}$ where U_(M) is an RMS value of a line-to-line motor voltage.
 18. The method of claim 10, wherein the common mode voltage is selected such that, for a maximum value for a line-to-ground voltage across terminals of a motor designed for operating directly off a sinusoidal power supply system, the following condition is met: ${\hat{u}}_{LEsystem} = {\frac{\sqrt{2}}{\sqrt{3}}U_{M}}$ where U_(M) is an RMS value of a line-to-line motor voltage. 